On the Deformation of the Circumflex Coronary Artery During Inflation Tests at Constant Length
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Transcript of On the Deformation of the Circumflex Coronary Artery During Inflation Tests at Constant Length
On the Deformation of the Circumflex Coronary ArteryDuring Inflation Tests at Constant Length
U. Saravanan & S. Baek & K.R. Rajagopal &
J.D. Humphrey
Received: 7 February 2006 /Accepted: 4 May 2006 / Published online: 13 July 2006# Society for Experimental Mechanics 2006
Abstract Here we investigate whether the deforma-
tion observed in an experiment in which the porcine
circumflex coronary artery is subjected to inflation at
constant length included in the class, r¼rðRÞ, �¼Q,
z¼LZ. We find that this is not the case and discuss its
implications in the study of the mechanics of this
artery. Moreover, we identify and quantify the uncer-
tainty in the value of the invariants of the left Cauchy–
Green tensor inferred from the 2D motion of markers
affixed to the surface of the test specimen, and suggest
that 3D tracking of markers is needed due to inherent
bending and twisting induced by pressurization in
vitro.
Keywords Coronary artery . Inflation tests . Non-
axisymmetric deformation . 2D marker tracking .
Calibration
Introduction
The stress experienced by cells in the arterial wall
modulates the structural and functional characteristics
[1–5]. Hence, we must quantify their transmural stress
distribution so that the role of mechanical factors can
be understood in arterial physiology and pathophysi-
ology. Towards this end, the present study aims to
glean information regarding the deformation field of
the circumflex coronary artery inflated at constant
length in vitro.
Coronary artery disease is a leading cause of
mortality in the western world, yet few studies address
the mechanics of these arteries (see [6]). Most of the
available data [7–14] concern the realized outer
diameter, for a given radial component of the normal
stress at the inner surface of the artery (usually
referred to as the lumenal pressure), when length is
held fixed during in vitro experiments or in unknown
conditions1 in vivo. These measurements alone are
inadequate to characterize the inhomogeneity or
anisotropy of the artery, for many constitutive pre-
scriptions can reasonably fit the available experimental
data.2 Hence, there is a need for additional informa-
tion about the deformation field.
One can consider the possible inhomogeneity and
anisotropy by observing the deformation of markers
placed on the surface of the circumflex artery. From this,
we could obtain the circumferential and axial variations
of the surface deformation field. Of course, this too is
insufficient for obtaining robust 3D constitutive relations,
which would also require information about the trans-
Experimental Mechanics (2006) 46: 647–656
DOI 10.1007/s11340-006-9036-2
U. Saravanan (*)Department of Civil Engineering, IIT-Madras Chennai,Tamil Nadu 600036, Indiae-mail: [email protected]
S. Baek : J.D. HumphreyDepartment of Biomechanical Engineering,Texas A&M University,College Station TX-77845-3120, USA
K.R. RajagopalDepartment of Mechanical Engineering,Texas A&M University,College Station TX-77845-3123, USA
2 This is the case for other arteries as well. Also, while Laplace’slaw is reasonable to estimate the circumferential stresses forhomogeneous, isotropic, thin walled bodies, it is not forinhomogeneous, anisotropic bodies and for those bodies whichhave internal stresses even when free of traction on theboundary.
1 Perivascular tissue may allow small changes in length and limitthe amount of distension, due to the generation of a radialcomponent of the normal stress at the outer surface.
SEM
mural variation of the deformation field (to infer the
radial inhomogeneity). Further, one expects that anisot-
ropy and the stress field in the boundary traction free
reference configuration of the artery will be revealed by
studying the eigen-directions of the left Cauchy–Green
stretch tensor in conjunction with the estimated eigen-
directions of the Cauchy stress tensor, and inhomogeneity
by the non-uniformity of the principal invariants of the
right Cauchy–Green stretch tensor evaluated over theo-
retically predetermined surfaces. Herein we focus on
invariants rather than eigen-directions and address the
possible existence of inhomogeneity.
Of course, one can glean information about inho-
mogeneity by performing experiments on the intact
artery and repeating the same after separating the
media and adventitia, as done by Lu et al. [15] for
coronary arteries and by Von Maltzahn et al. [16] for
carotid arteries. Apart from difficulties in dissection,
this will alter the self equilibrating stress field in the
boundary traction free reference configuration of the
body. Hence, any observed changes in mechanical
response would be due in part to the altered stress field
in the configuration chosen as reference and different
material properties of the media and adventitia.
Therefore, there is an advantage to infer the stress
field in the reference configuration and inhomogeneity
within the context of a boundary value problem on
intact arteries rather than inferring them from destruc-
tive experiments. Since different stress fields in the
reference configuration and inhomogeneities would
theoretically result in different deformation fields, we
seek to deduce them by obtaining information regard-
ing the deformation. However, many distinct stress
fields in the reference configuration and inhomogene-
ities could result in deformation fields that are too
close to be resolved experimentally due to the
uncertainty associated with the estimated deformation
field, leading to non-uniqueness with regard to the
inverse problem at hand. Hence, we also study the
experimental uncertainty as well.
Here we illustrate our ideas by studying the
response of porcine circumflex coronary arteries sub-
jected to inflation at constant length. It is commonly
assumed that the deformation of arteries subjected in
vitro to inflation at constant length is given by
r ¼ rðRÞ; � ¼ Q; z ¼ LZ; ð1Þ
where ðR;Q;ZÞ denotes the cylindrical polar coordi-
nates of a typical material point in a reference
configuration and ðr; �; zÞ denotes the cylindrical polar
coordinates of a typical material point in the current
configuration. In general, such a deformation is
possible in annular right circular cylinders only when
the body is at most radially inhomogeneous and the
stress field in the reference configuration could vary at
most radially. Otherwise, the equilibrium equations
cannot be satisfied. This means that if the observed
deformation is of the form (1), then the two-layered
annular right circular cylinder approximation of the
artery can be accommodated. Here we investigate
whether a deformation of the form (1) is possible in a
circumflex coronary artery that is inflated and held at
constant length, in vitro. In vivo, it has been shown by
Pao et al. [17] that coronary arteries are subjected to
axial extension and torsion in addition to the longitu-
dinal shear at the inner surface of the artery due to the
flowing blood and inflation due to the blood pressure;
this complexity arises, in part, because of changes in
shape and size of the heart during the cardiac cycle. In
vitro we also find that the artery bends and twists on
inflating when holding it at constant length; this
implies that the deformation is not of the form (1). It
is pertinent to note that Draney et al. [18], studying
porcine aortic wall motion in vivo using cine phase
contrast MRI, report circumferentially non-uniform
deformation. Thus, it appears that in many arteries the
deformation might not be of the form (1), which has
profound implications in the study of the mechanics of
these arteries which we discuss in some detail.
Materials and Methods
Experimental System
A computer controlled system, originally designed and
built to test embryonic chick hearts subjected to low
pressures [19], was adapted to test porcine circumflex
coronary arteries. The overall system consists of three
main subsystems (Fig. 1).
We employ a video-based system that allows 2D
tracking of up to 12 surface markers. This system
consists of a microscope (Olympus SZ60) with an
auxiliary viewing port (SZ-PT), a charged couple
device (CCD) camera (Javelin JE-7442), a VCR (Sony
SVT-S3100), two B&W monitors (Sony SSM-171 for
specimen preparation and a Panasonic TR-930B for
visualizing the on-line tracking of fiducial markers),
and a video frame grabber board (Data Translation
DT-2853SQ) that captures 8 bit gray scale images as
512� 512 pixel arrays. Markers are tracked online at
30 Hz using the correlation-based algorithm reported
in Downs et al. [20]. To maintain the focus of the
markers on the surface of the artery during Bextreme^deformations, a manually controlled focussing mecha-
nism translates the microscope optics vertically. This
648 Exp Mech (2006) 46: 647–656
SEM
was achieved by replacing the rack and pinion
microscope stand with a motorized vertical translation
stage (Newport Corporation 426 and CMA-25CC 861
controller) mounted on a damped mounting rod
(Thorlabs DP14).
Second, the cannulated specimen is held and loaded
by means of a mounting system, so that the artery is
submerged in the test chamber containing a physio-
logic solution. The specimen can be axially stretched
using paired computer controlled actuators (Newport
Corp.) through precision x–y–z stages that adjust the
position of the specimen within the video field of view.
The x–y–z stages also maintain the length of the artery
during inflation. One end of the specimen is attached
to a computer controlled syringe pump (World Preci-
sion Instruments SP210iw) and the other end to a
pressure transducer (Sensotec) and load cell (Senso-
tec), as shown in Fig. 1. The syringe pump, fitted with a
3 cc syringe (Hamilton 1705TLL), is controlled by the
computer via ASCII commands that allows cyclic
pressurization tests over a wide range of infusion rates.
The pressure transducer has a sensing range from 0 to
258 mmHg, with a factory reported accuracy of
0.26 mmHg. The axial load cell has a sensing range
from 0 to 250 g with a reported accuracy of 0.25 g. The
pressure transducer and the load cell are sampled via a
12-bit analog to digital (A/D) board (Data Translation
DT2831) in the computer.
Third, the experiments and data collection (video,
axial load and lumenal pressure) are controlled by
keyboard commands via a custom C code running on
an Intel Pentium II computer (Compaq Deskpro,
RAM reduced to 8 MB to accommodate the online
tracking algorithm). The stored data are analyzed
offline using a custom matlab code.
The pressure transducer was calibrated using a
sphygmomanometer and the load cell using standard
weights. The video system was not calibrated because
we were interested only in the dimensionless gradient
of the deformation.
Computation of the Deformation Gradient
We estimate a smooth deformation field from posi-
tions of Fn_ markers in the reference and current
configuration and then compute the gradient of the
deformation field. In general, it is not possible to
experimentally determine the exact deformation field
by tracking Fn_ markers, we can at most get a reasonable
approximation of the deformation field and its gradient
locally. However, we can verify if the observed defor-
mation field is consistent with that theoretically pre-
dicted. Towards this end we shall see that if the artery
were to deform as given in equation (1), then it suffices
to assume that the deformation field on the surface of
the specimen in a centered gage length is given by
x ¼ ax1X þ ax
2Z þ ax3; z ¼ az
1X þ az2Z þ az
3; ð2Þ
where axi and az
i are constants and ðx; zÞ denotes the
2D coordinates of the markers in the current configu-
ration and ðX;ZÞ the corresponding coordinates in a
reference configuration. Knowing the location of three
markers in the current and reference configurations,
we can obtain ðaxi Þ
c and ðazi Þ
c, with the value of axi and
Fig. 1 Schematic of theexperimental setup
Exp Mech (2006) 46: 647–656 649
SEM
azi corresponding to the cth choice of three markers,
from solving the linear equations
X1 Z1 1
X2 Z2 1
X3 Z3 1
0B@
1CAðax
1Þc
ðax2Þ
c
ðax3Þ
c
8><>:
9>=>;¼
x1
x2
x3
8><>:
9>=>;;
X1 Z1 1
X2 Z2 1
X3 Z3 1
0B@
1CAðaz
1Þc
ðaz2Þ
c
ðaz3Þ
c
8><>:
9>=>;¼
z1
z2
z3
8><>:
9>=>;;
ð3Þ
where Xi and Zi are coordinates in the reference
configuration of the ith marker that belongs to the
three markers that have been selected and xi and zi are
the coordinates of the same ith marker in the current
configuration. It is then straightforward to see that the
invariants, trðC2DÞ and detðC2DÞ, are given by
ðI2D1 Þ
c ¼ ðax1Þ
c2 þ ðax2Þ
c2 þ ðaz1Þ
c2 þ ðaz2Þ
c2;
ðI2D3 Þ
c ¼ ½ðax1Þ
cðaz2Þ
c � ðax2Þ
cðaz1Þ
c�2;ð4Þ
respectively, where, C¼FtF is the right Cauchy-Green
stretch tensor and F is the deformation gradient. Thus,
we find ðI2D1 Þ
c and ðI2D3 Þ
c corresponding to the cth
choice of three markers. Figure 2 shows a typical
selection of 12 sets of three markers where the markers
are at the vertices of each triangle and are denoted by
arabic numerals. Here we choose different sets of
three markers such that the triangles formed with
these markers as vertices have no overlapping areas.
Sometimes, one or two of the markers would wash off,
in which case the triangles were formed with remaining
markers still ensuring no overlap of the areas.
A study on the quality of approximation
Next, let us study in some detail the consequences of
approximating the deformation (1) using a linear
polynomial, (2). Let ðRo;Q1;Z1Þ, ðRo;Q2;Z2Þ, ðRo;Q3;
Z3Þ denote the cylindrical polar coordinates of three
markers in the reference configuration and ðro; �1; z1Þ,ðro; �2; z2Þ, ðro; �3; z3Þ the cylindrical polar coordinates
of the same markers in the current configuration. Now,
equation (3) becomes
Ro cosðQ1Þ þ xo Z1 1
Ro cosðQ2Þ þ xo Z2 1
Ro cosðQ3Þ þ xo Z3 1
0B@
1CA
ax1
ax2
ax3
8><>:
9>=>;¼
ro cosð�1Þ þ xo
ro cosð�2Þ þ xo
ro cosð�3Þ þ xo
8><>:
9>=>;;
Ro cosðQ1Þ þ xo Z1 1
Ro cosðQ2Þ þ xo Z2 1
Ro cosðQ3Þ þ xo Z3 1
0B@
1CA
az1
az2
az3
8><>:
9>=>;¼
z1
z2
z3
8><>:
9>=>;;
ð5Þ
where ro¼rðRoÞ and xo shifts the origin from the axis
of the annular cylinder to some point outside the
cylinder, which happens when local coordinates of the
frame grabber board are used. Solving the above
equations for axi and az
i and using �¼Q and z¼LZ,
we obtain ax1¼ro=Ro, ax
2¼0, ax3¼ðRo � roÞxo=Ro, az
1¼az
3¼0 and az2¼L. Thus, the value of the constants a
ji are
independent of the choice of the three markers selected,
as long as they are on the surface of the artery. The
values of
I2D1 ¼ ro
Ro
� �2
þL2 and I2D3 ¼ ro
RoL
� �2
; ð6Þ
are constant when inferred from tracking markers on
the surface of the artery, if assumed to be a right
circular annular cylinder and the actual deformation is
given by equation (1). It is this constancy of the
principal invariants that we propose to test. Also, we
have verified that equation (2) is sufficient for com-
puting the deformation gradient when the actual
deformation is given by equation (1).
Sample Preparation
Animal care in this study conformed to the guidelines
of the University Laboratory Animal Care Committee,
Texas A&M University. Hearts of micro-mini pigs
(Panapinto Micro Minipigs; Mansonville, CO) used in
another (approved) study were harvested and trans-
ported in ice-cold normal saline. Two to four cm long
segments of the circumflex artery, from its origin at the
left coronary artery, were dissected (see Fig. 3) and its
side branches were ligated using 2-0 or 3-0 nylon
150 200 250 300 350 400
0
50
100
150
200
250
Z (Pixel)
X (
Pix
el) I
II
III
IV
V
VI
VII
VIII
IX X
XI XII
1
2
3
4
5
6
7
8
9
10
11
12
Fig. 2 Selection of triangles (I–XII) in the reference configura-tion to compute the deformation field by tracking 12 markers (1–12) using equation (2)
650 Exp Mech (2006) 46: 647–656
SEM
braided sutures, depending on the size of the branches.
Care was exercised to ensure that minimal perivascular
tissue was attached to the ligatures (see Fig. 4). The
excised circumflex artery was mounted on two stainless
steel cannulae, with outer diameters nearly equaling
the inner diameter of the circumflex artery and care
being exercised to ensure that the artery did not twist.
Then, the vessel was held fixed at its unloaded length,
denoted Lo. It should be pointed that the in vivo
length of the circumflex changes with the inflation and
deflation of the heart and hence is not well defined.
Subsequently 100 mm diameter black spheres (Interac-
tive Medical Technologies) made of polystyrene
divinylbenzene were placed on the surface of the
artery using fine tipped forceps and glued (Perma-
bond) using a glass micropipet (WPI PG52150-4)
which was formed using a pipet puller (World Preci-
sion Instruments PUL-1) and by grinding it down to
the desired diameter of 50 mm. The location of the
markers was approximately at the center of the artery
and not near the ligations, when possible.
Protocols
On each of 30 specimens the following protocols were
performed:
1. The locations of the markers on the adventitia, in a
configuration free of boundary traction, were
recorded under quiescent conditions and defined
the native reference configuration. The invariants
I2D1 and I2D
3 , were computed using this as the
reference configuration.
2. The specimen was translated along the x direction
using the actuators in the precision x–y–z stages
and the motion of the markers recorded. This
protocol was performed to estimate the error in the
video tracking system.
3. The microscope was translated vertically using the
motorized actuator described before, and the
motion of the markers tracked. This protocol was
performed to estimate the error in the video
tracking system due to changing focus.
4. The artery was cyclically inflated and deflated from
1 mm Hg to 120 mm Hg for five cycles at constant
length in a normal saline bath (154 mM NaCl) by
infusing and withdrawing normal saline at 15ml=s.
The response was called native because the artery
was assumed to be in the native state i.e., isolated
from natural or artificial hormonal and neural
stimuli.
Other protocols were performed in many speci-
mens, including tests in solutions with high potassium
concentration to activate the smooth muscle followed
by tests in low calcium solutions to deactivate the
smooth muscle. Because the key finding on inhomo-
geneity was observed independent of the test solution,
the normal saline results are given here. See Saravanan
[21] for further details and results.
Results
Uncertainty Analysis
Any experimental measurement has some uncertainty
associated with it and it is necessary to estimate the
level of uncertainty. Towards this end, we start with
examining the error associated with determining the
location of the centroid of each marker. That is, the
determined location of a marker will usually be within
only a certain number of pixels of the actual location
thereby inducing an error. Further, the location of a
marker can only change discretely during tracking, as
opposed to continuous variations in reality. To get an
estimate of these errors, three protocols elaborated
above were used.
First, the initial location of markers was recorded
over 10 seconds in the reference configuration. The
Fig. 3 Schematic of the location from where the circumflexcoronary artery is dissected. LAD stands for left anteriordescending artery
Fig. 4 A dissected circumflex coronary artery. Note the naturalcurvatures
Exp Mech (2006) 46: 647–656 651
SEM
mean of all the repeated recordings was taken as the
location of a marker. Now, for the locations of the
markers in the current configuration, we used the same
readings obtained while recording the initial location
of the markers. Hence, ideally ðI2D1 Þ
c¼ 2 and ðI2D3 Þ
c¼ 1
and any deviation from these values signifies an error.
The deviation occurs because the centroids are deter-
mined within an accuracy of �a pixels due to inherent
noise in the system. When the deformation was
approximated by a linear polynomial (2), which was
determined using three markers, ðI2D1 Þ
c�2 and
ðI2D3 Þ
c�1 varied by as much as �0:02. This error was
sensitive to the number of readings, Fb_, over which the
averaged location of the markers was computed in the
current configuration, the polynomial used to approx-
imate the deformation, and the particular selection of
the markers. This error decreased as the number of
readings over which the marker location was averaged
increased, and decreased as the area subtended by the
triplets increased. However, as the area subtended by
the markers increased, the quality of the approximation
of the deformation and its gradient by linear polyno-
mial decreased. Hence, a balance has to be maintained.
Second, the repeated recording of an initial static
configuration of the markers was used to find the
location of the markers in the reference configuration
and protocol 2, in which the markers were translated
as a rigid body along the x direction, was used for the
location of the markers in the current configuration.
As before ideally, ðI2D1 Þ
c¼ 2, ðI2D3 Þ
c¼ 1. A represen-
tative plot of these errors for ðI2D1 Þ
c � 2 is shown in
Fig. 5(a) when the deformation was approximated by a
linear polynomial, determined using three markers,
and when the markers were manually translated by 300
pixels along the x direction in 18 seconds.3 Figure 5(b)
plots the histogram from the data in Fig. 5(a). Similar
plots were obtained for ðI2D3 Þ
c � 1 (not shown). While
the error increased with decreases in the area sub-
tended by the triplet of three markers, it initially
decreased but then increased with increasing number
of readings over which the averaged location of the
markers was computed. Hence, there exists an optimal
number of readings averaging over which the error is a
minimum. From this study, we found that averaging
over ten readings of the marker location appears to be
optimal in finding the true mean.
Finally, the third protocol was used to estimate the
error introduced due to changing focus. The reference
configuration was inferred as before, but the current
configuration of the markers was inferred from record-
ings in protocol-3. Again, ideally ðI2D1 Þ
c¼ 2 and
ðI2D3 Þ
c¼ 1. When the deformation was approximated
by a linear polynomial, using three markers, and when
the microscope was translated by �1250mm, the
estimated value of ðI2D1 Þ
c�2 and ðI2D3 Þ
c�1 changed by
as much as �0:06. This error was sensitive to the same
variables described above and changed in the same
manner as illustrated in Fig. 5. From these studies it
was concluded that the error in the estimated invari-
ants is �0:06.
Next, we examined the gross error associated with
2D tracking of the markers. First, we note that
markers placed on the surface of an artery do not lie
on a plane. Further, if the deformation is not of the
form (1), significant systematic errors can be intro-
duced due to the limitation of 2D tracking. To
estimate the error, a numerical simulation was per-
0 50 100 150
−0.05
0
0.05
Non dimensional time
(I12D
)c 2
(a)
0.05 0 0.050
100
200
300
400
500
µ = − 0.003
σ = 0.017
(I12D)c − 2
Fre
quen
cy
(b)
−
1 2 42 4 52 3 53 5 64 5 75 7 85 6 86 8 97 8 108 10 11
− − −−−−
− − −−−−
− − −−−−
− − −−−−
− − −
8 9 11− − −9 11 12− − −
− − −
Fig. 5 Plot of ðI2D1 Þ
c�2 as a (a) time series (b) histogram while
translating the artery along the x direction as a rigid body. Each
symbol type in panel (a) denotes a different triplet of markers
3 Typically, while inflating the artery the markers translate 300pixels along the x direction in 32 seconds
652 Exp Mech (2006) 46: 647–656
SEM
formed. For a rigid body rotation about its axis, i.e.,
the artery was assumed to deform as
r ¼ R; � ¼ � þ Q; z ¼ Z; ð7Þ
and the value of the invariants was computed theoret-
ically under the assumption that the markers were
tracked in 2D using equation (5). Figure 6 reveals that
the value of the invariants are far from their expected
values, ðI2D1 Þ
c¼ 2 and ðI2D3 Þ
c¼ 1. Thus, while this ex-
perimental set-up is ideal if the artery deforms as given
by equation (1), caution has to be exercised on inter-
preting the data when the deformation differs.
Next, we turn our focus to errors that are more
difficult to quantify. Some twist could be introduced
inadvertently while mounting the artery, and the effect
of this on the deformation of the artery while inflating
requires quantification. Towards this end, holding one
end fixed, the other end of the artery was rotated
manually so that the twist per unit length W was
approximately 1 deg/mm. Figure 7 depicts ðI2D1 Þ
c for
combined inflation at a fixed extension and twist of the
artery; note that the variation of ðI2D3 Þ
c is similar to
that of ðI2D1 Þ
c. In the same figures the response of the
artery when there was no twist is presented for
comparison. The presence of twist not only increased
the value of the invariants for a given pressure, as it
should, the variation was also larger when evaluated at
different locations on the surface of the artery. This
dependence of the invariants on the location on the
outer surface at which they were evaluated is expected
because twisting causes out of plane deformation of
the markers, which the 2D tracking system was unable
to capture correctly. Figure 8 depicts the invariants
when the artery was inflated by applying a pressure at
its inner surface from the twisted reference configura-
tion. In other words, the only difference between
Fig. 8 and Fig. 7(b) is the reference configuration used
to compute the value of the invariants. This is the
situation when the artery is mounted incorrectly, i.e.,
with a twist. Comparing Fig. 8 with Fig. 7(a), we find
that while the magnitude of the invariants were com-
parable when one accounts for the axial extension, their
variation with the choice of the markers was different
for lower pressures. This is because the invariants are
constrained to be ðI2D1 Þ
c¼ 2 and ðI2D3 Þ
c¼ 1 in the latter
case when the pressure is 0.
Finally, gluing markers onto the surface of the
artery introduces some error in the measured defor-
mation. The motion of the markers would also be
Fig. 6 Theoretically computed plots of I2D1 �2 and I2D
3 �1 when
the deformation of the artery is given by equation (7) for various
values of �. Note that both I2D1 �2 and I2D
3 �1 are close to each
other. The X and Z values listed in the figure gives the initial
coordinates of the markers constituting the triplet
0 20 400
0.5
1
1.5
2
β (deg)
Inva
riant
s
X = [157 152 110]
Z = [200 160 194]
(I12D)c − 2
(I32D)c − 1
0 20 40 60 80 100 120
0
0.5
1
1.5
Pressure (mm Hg)
(I12D
)c − 2
1 2 42 4 52 3 53 5 64 5 75 7 85 6 86 8 117 8 98 9 108 10 11
(a)
0 20 40 60 80 100 120
0
0.5
1
1.5
Pressure (mm Hg)
(I12D
)c 2
(b)
−
− − −−−−
− − −−−−
− − −−−−
− − −−−−
− − −−−−
− − −
Fig. 7 Plot of ðI2D1 Þ
c�2 when L¼1:1aW¼0bW¼1deg=mm for a
29 mm long vessel and inflating the artery to 120 mm Hg
Exp Mech (2006) 46: 647–656 653
SEM
influenced by the ligations of the side branches. These
errors are not quantified here, as they are difficult to
assess. However, these can be viewed as perturbations
that are a necessary adjunct of the experimental
measurements.
Results from Inflation Tests
Figure 9 displays how the pressure varied with the
invariants computed with respect to the native refer-
ence configuration corresponding to the 4th cycle of
loading and unloading. Contrary to expectation, we
see from the figure that the invariants seem to vary
spatially. The spatial variation of the invariants is far
more than can be accounted for by the error in the
location of their centroid, which was estimated to
cause a deviation of �0:06 in the value of the
invariants. Hence, the deformation of the artery
subjected to inflation at constant length is not given
by equation (1). The same conclusion was reached for
all the specimens tested. Although not shown, the
variability in the value of the invariants depended on
the vascular smooth muscle tone and the axial stretch
ratio at which the vessel was held constant (see
Saravanan [21]). In fact, during the experiments one
could observe bending and twisting of the artery when
inflated, at a constant length, which we hypothesize to
be responsible for the observed variation in the value
of the invariants with the choice of the markers.
It is pertinent to note that Han and Fung [22], while
investigating the pre-strain in porcine aorta by intro-
ducing a radial cut on a transverse section, also report
local circumferential variation of the components of
the pre-strain apart from the radial variation (see their
Fig. 3), that is for small variations in the circumferen-
tial and radial location. However, globally the circum-
ferential variation was not statistically significant.4 In a
pilot study, we found that the deformation field varied
significantly for diametrically opposite locations during
inflation of the artery at constant length (see Fig. 10).
These observations suggest further that the deforma-
tion of the circumflex coronary artery inflated at
constant length does not correspond to equation (1).
Fig. 9 Plot of ðI2D1 Þ
c�2 for (a) specimen-1 (b) specimen-2 com-
puted for various marker sets while inflating the porcine circumflex
artery, in the native state at constant length, Lo. A similar plot was
obtained for ðI2D3 Þ
c�1 in the case of both specimens (not shown).
Symbols are the same as in Fig. 7
0 20 40 60 80 100 120
0
0.5
1
1.5
Pressure (mm Hg)
(I12D
)c 2
(a)
0 20 40 60 80 100 120
0
0.5
1
1.5
Pressure (mm Hg)
(I12D
)c 2
(b)
−−
0 20 40 60 80 100 120
0
0.5
1
1.5
Pressure (mm Hg)
(I12D
)c − 2
Fig. 8 Plot of ðI2D1 Þ
c�2 when L¼1, W¼1deg=mm and inflating
the artery to 120 mm Hg. A similar plot was obtained for ðI2D3 Þ
c�1(not shown). Symbols are the same as in Fig. 7
4 This just means that the deformation is a non-linear function ofthe radial location contrary to the assumption made whilecomputing the strain from the location of the markers in thecurrent and reference configuration. In fact, the theoreticallydetermined deformation field, as reported by them, is a non-linear function of FR_, the radial location.
654 Exp Mech (2006) 46: 647–656
SEM
Discussion
Unlike the common carotid or basilar artery, the
excised circumflex coronary artery is not straight (see
Fig. 4): it has a natural curvature and it tapers, in
addition to having many branches that need to be
ligated. These ligations and the geometry of the vessel
can result in the deformation not being of the form (1).
Fosdick [23] has shown that the deformation of the
form5
r ¼ f ðR; tÞ; � ¼ Q; z ¼ �Z; ð8Þ
is possible in all homogeneous, incompressible, isotro-
pic bodies when inertial effects are taken into account.
This result can be extended to include all radially
inhomogeneous, incompressible, isotropic bodies. For
certain classes of stored energy function that seem to
describe arteries reasonably well, Humphrey and Na
[24] have shown that the difference between the quasi-
static and the dynamic solution is small when the rate
of change of the radial component of the normal stress
at the inner surface coincides with the observed
variation of the blood pressure. In our study, the rate
of change of the radial component of the normal stress
was much smaller6 than that of the rate of change in
the blood pressure. Hence, it seems unlikely that the
observed difference in the deformation could be
explained by including inertial effects.
We found that when a small segment of the
circumflex coronary artery obtained from the proximal
portion (i.e., near the aorta) was cut radially, the
opening angle (as defined in Choung and Fung [25])
was greater than that obtained from the distal portion,
i.e., the opening angle changes significantly along the
axial direction over a 20 to 40 mm length of the
circumflex coronary artery.7 This empirical observa-
tion suggests that the stress field in the reference
configuration varies axially as well as radially.
An anisotropic body cannot support an arbitrary
stress field in the reference configuration. Coleman
and Noll [27] determined the states of stresses that are
compatible with the anisotropy of the body, within the
context of elasticity. Hoger [28] determined restric-
tions on the residually stressed field that, in addition to
being consistent with the anisotropy of the body,
satisfies the equilibrium equations and the appropriate
traction boundary condition. The fact that the body
under consideration is anisotropic and inhomogeneous
and has to satisfy the equations of equilibrium implies
that the artery ought to bend and twist when subjected
to the type of loadings that were considered in this
paper. Of course, either the anisotropy or inhomoge-
neity or both might be responsible for the observed
deformation.
It has been conjectured that bending and twisting
are responsible for coronary arteries being prone to
atherosclerosis [29–31]. Hence, it becomes necessary to
investigate the cause for bending and twisting of the
artery. This would at the least require the capability to
track the surface markers in 3D, to measure the torque
that needs to be applied while inflating the vessel to
maintain a given angle of twist, and to investigate the
orientation of the collagen, elastin, and vascular
smooth muscle cells. Tracking surface markers in 3D
can be accomplished with two cameras (i.e., a biplane
video system) and the torque can be measured with a
standard transducer. Although, pressure diameter
studies provide some information we conclude, that
future Binflation-extension^ experiments on arteries
having natural out of plane curvatures be augmented
with these experimental capabilities and that histology
be performed regionally as a function of axial and
circumferential location, not just radial.
Acknowledgments This work was supported, in part, by NIHgrant R01-HL64372. We thank Dr. J.J. Hu for the artwork of theexperimental setup.
5 ðR;Q;ZÞ are the cylindrical polar coordinates of a typical pointin the reference configuration and ðr; �; zÞ are the cylindricalpolar coordinates of a typical point in the current configuration.6 In the present case, the pressure increased approximately atthe rate of 1 mmHg/s. In the experiments we maintained theinfusion and withdrawal rate to be constant and not the pressure. 7 The same was shown for rat aorta by Liu and Fung [26].
0 20 40 60 80 100 120
0
0.5
1
1.5
Pressure (mm Hg)
(I12D
) c −
2Std. Err at loc 1Mean at loc 1Std. Err. at loc 2Mean at loc 2
−−
−−
Fig. 10 Plot of ðI2D1 Þ
c�2 inferred from diametrically opposite
locations while inflating the circumflex artery holding it at a constant
length, 1:1Lo. A similar plot was obtained for ðI2D3 Þ
c�1 (not shown)
Exp Mech (2006) 46: 647–656 655
SEM
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